Alloys for hardbanding weld overlays

ABSTRACT

Disclosed herein are iron-based alloys having a microstructure comprising a fine-grained ferritic matrix and having a 60+ Rockwell C surface, wherein the ferritic matrix comprises &lt;10 μm carbide precipitates. Also disclosed are methods of welding comprising forming a crack free hardbanding weld overlay coating with such an iron-based alloy. Also disclosed are families of alloys capable of forming crack-free weld overlays after multiple welding passes.

INCORPORATION BY REFERENCE TO ANY PRIORITY APPLICATIONS

Any and all applications for which a foreign or domestic priority claim is identified in the Application Data Sheet as filed with the present application are hereby incorporated by reference under 37 CFR 1.57.

TECHNICAL FIELD

The present invention relates generally to metallurgy. More particularly, some embodiments relate to: amorphous, nanocrystalline, or microcystalline metals; and weld overlay materials.

DESCRIPTION OF THE RELATED ART

Amorphous metallic materials made of multiple components with a non-crystalline structure are also known as “metallic glass” materials. The materials often have different behaviors from corresponding metals with crystalline structures. Notably, an amorphous metallic material is usually stronger than a crystalline alloy of the same or similar composition. Bulk metallic glasses are a specific type of amorphous materials or metallic glass made directly from the liquid state without any crystalline phase. Bulk metallic glasses typically exhibit slow critical cooling rates, e.g., less than 100 K/s, high material strength and high resistance to corrosion. Bulk metallic glasses may be produced by various processes, e.g., rapid solidification of molten alloys at a rate that the atoms of the multiple components do not have sufficient time to align and form crystalline structures. Alloys with high amorphous formability can be cooled at slower rates and thus be made into larger volumes and can be produced using common industrial practices such as thermal spray processing or welding. The determination of an amorphous material is commonly made using X-ray diffractometry. Amorphous materials lack translational symmetry, and thus produce X-ray diffraction spectra composed of a single broad hump as opposed to the sharp peaks defined over a narrow diffraction angle range typical to crystalline materials.

The formation of metallic glasses is very complex as compared to conventional crystalline materials, and thus modeling efforts designed to understand and predict production of metallic glasses are not very accurate. Many modeling criteria have been developed to predict certain aspects of metallic glass design. These models typically fail to include specific quantifiable components and therefore fail to provide concrete metallic glass formation ranges. As a result, metallic glasses are developed primarily through a trial and error experimental process, where many alloys must be produced and evaluated before a metallic glass composition is discovered.

Despite the many advantageous properties of metallic glasses, it is often useful to contain a level of crystalline in the material ranging from a small fraction to completely crystalline. Nanocrystalline or fine-scale grained materials are known to contain higher hardness and strength than equivalent larger grained materials. Metallic glasses are known to form nanocrystalline precipitates when cooled a slower rate than their glass forming ability requires. Even slower cooling produces complete crystallinity ranging from nanometer sized grains and up. In general, materials which form metallic glasses have slower crystallization kinetics and will thus form smaller grain sized than common materials processed under the same conditions. In addition controlling the rate of cooling, it is often possible to dictate the crystallinity fraction and grain size of a material though compositional control. By altering the composition from its optimum glass forming concentration, the precipitation of a particular crystalline phase can be encouraged under appropriate processing conditions. This technique has been used to increase ductility in metallic glasses.

Most materials, even those capable of forming completely amorphous structures under thermal spray processing, do not have slow enough crystallization kinetics to form an amorphous material when welded. Nevertheless, the crystallization kinetics are such that a fine-scale grain structure is likely to form.

Most hardfacing materials, especially when dealing with weld overlays capable of exceeding 60 Rockwell C hardness, suffer from cracking during the weld process as well as poor toughness. In addition to other problems, this cracking limits such a materials use in any application where impact occurs. Accordingly, the durability of hardfacing weld overlays can be substantial improved by reducing the potential for cracking and increasing the overall toughness of the weld.

Using tungsten carbide (“WC”) as a hard particle reinforcement in the weld overlay technique is another typical method of hardfacing. This technique involves pouring WC into the molten weld bead as the hardfacing material is being welded onto the substrate. In many applications this technique offers a very good hardfacing layer, however it is difficult to apply a hardfacing layer of this type using a hard material as the matrix for the WC particles, particularly when cracking in the hardfacing layer is not desirable. Extreme wear applications often demand improved wear performance beyond that which can be offered using a ductile matrix with WC particles, because the matrix itself is likely to wear away at an accelerated rate leaving the hard particles exposed to shatter or pull out from the surface. Under conditions of extreme impact as well as wear it is important to eliminate cracking in the weld bead.

Hardbanding is a technique used to protect the drill stem during operation in oil and gas drilling. The hardbanding is a weld overlay made onto a round tool joint, typically 6″ in diameter, which is applied in the field. The hardbanding overlay is designed to be a hard wear resistant alloy which centers the drill stem within the casing, as well as protects the drill stem from wearing itself away on the casing.

BRIEF SUMMARY OF EMBODIMENTS OF THE INVENTION

According to certain aspects of the present disclosure, weld overlay materials are disclosed. In some embodiments, one or more materials of the present disclosure can be used as a superior weld overlay material for the protection of tool joints in oil and gas drilling operations. In some embodiments, one or more materials of the present disclosure can be used for other overlay hardfacing applications.

According to certain aspects of the present disclosure, an iron-based alloy is provided. The alloy can have a microstructure comprising a fine-grained ferritic matrix. The alloy can have a 60+ Rockwell C surface. The ferritic matrix can comprise <10 μm Nb and W carbide precipitates.

According to certain aspects of the present disclosure, a method of welding is provided. The method can comprise forming a crack free hardbanding weld overlay coating with an iron-based alloy. The alloy can have a microstructure comprising a fine-grained ferritic matrix. The alloy can have a 60+ Rockwell C surface. The ferritic matrix can comprise <10 μm Nb and W carbide precipitates.

According to certain aspects of the present disclosure, a method of designing an alloy capable of forming a crack free hardbanding weld overlay is provided. The method can comprise the step of determining an amorphous forming epicenter composition. The method can further comprise the step of determining a variant composition having a predetermined change in constituent elements from the amorphous forming epicenter composition. The method can further comprise forming and analyzing an alloy having the variant composition.

Other features and aspects of the invention will become apparent from the following detailed description, taken in conjunction with the accompanying drawings, which illustrate, by way of example, the features in accordance with embodiments of the invention. The summary is not intended to limit the scope of the invention, which is defined solely by the claims attached hereto.

BRIEF DESCRIPTION OF THE DRAWINGS

The present invention, in accordance with one or more various embodiments, is described in detail with reference to the following figures. The drawings are provided for purposes of illustration only and merely depict typical or example embodiments of the invention. These drawings are provided to facilitate the reader's understanding of the invention and shall not be considered limiting of the breadth, scope, or applicability of the invention. It should be noted that for clarity and ease of illustration these drawings are not necessarily made to scale.

FIG. 1A is a table illustrating a variety of atomic radii for some elements that may serve as constituents of some embodiments of the invention.

FIGS. 1B-1I are graphs illustrating various characteristics of some embodiments of the invention.

FIG. 2 is an x-ray diffraction spectrum of an embodiment of the invention.

FIG. 3 is an x-ray diffraction spectrum of an embodiment of the invention.

FIG. 4 is an x-ray diffraction spectrum of an embodiment of the invention.

FIG. 5 is an x-ray diffraction spectrum of an embodiment of the invention.

FIG. 6 is a wear performance comparison between an embodiment of the invention and other materials.

FIG. 7 is a coefficient of friction comparison between an embodiment of the invention and other materials.

FIG. 8 is a galvanic potential comparison between an embodiment of the invention and another material.

FIG. 9 is a scanning electron microscope image of an embodiment of the invention.

FIG. 10 is a dry sand wear test comparison between an embodiment of invention and other materials.

FIG. 11 is a scanning electron microscope image of the results of a Vickers indentation test on an embodiment of the invention.

FIG. 12 is a scanning electron microscope image of an embodiment of the invention.

FIGS. 13A and 13B are scanning electron microscope images of an embodiment of the invention.

FIG. 14 is a scanning electron microscope image of an embodiment of the invention.

FIG. 15 is a scanning electron microscope image of an embodiment of the invention.

FIG. 16 is a scanning electron microscope image of an embodiment of the invention.

FIG. 17 is a scanning electron microscope image of an embodiment of the invention.

FIG. 18 is MIG weld bead of alloy on 4140 steel 6″ diameter pipe showing no cracking or cross-checking as measured using liquid dye penetrant.

FIG. 19 is a diagram depicting an alloy design process according to certain aspects of the present disclosure.

FIG. 20 is a graph illustrating an amorphous forming composition epicenter and an associated amorphous forming composition range according to certain aspects of the present disclosure.

FIG. 21 shows an exemplary arc melter that can be used to melt an homogeneous alloy ingot for solidification analysis.

FIG. 22 is a phase diagram that is used for predicting behavior of an alloy when specific alloying elements are either added or subtracted from an amorphous forming epicenter composition according to certain aspects of the present disclosure.

FIG. 23 is a diagram illustrating an exemplary alloy formation and analysis procedure.

FIG. 24 is a diagram depicting liquid composition versus cooling curves for various constituent compositions.

FIGS. 25A and 25B illustrate the result of welding the CFEXP-1 alloy onto a 6⅝″ 4137 steel tool joint with a single pass.

FIGS. 26A and 26B illustrate single passes of as-welded CFEXP-2 alloy on 6⅝″ 4137 steel tool joint.

FIG. 27 illustrates a single pass of as-welded CFEXP-5 alloy on 6⅝″ 4137 steel tool joint.

FIGS. 28A and 28B illustrate single passes of as-welded CFEXP-6 alloy on 6⅝″ 4137 steel tool joint.

FIGS. 29A and 29B illustrate as-welded CFEXP-11a on 6⅝″ 4137 steel tool joint.

FIGS. 30A and 30B illustrate as-welded CFEXP-12 alloy on 6⅝″ 4137 steel tool joint.

FIGS. 31A and 31B illustrate as welded CFEXP-13 alloy on 6⅝″ 4137 steel tool joint.

FIGS. 32A-C illustrate as-welded CFEXP-14 alloy on 6⅝″ 4137 steel tool joint.

FIG. 33 illustrates as-welded CFEXP-15 alloy on 6⅝″ 4137 steel tool joint indicating no cracks.

FIGS. 34A and 34B illustrate the results of welding with CFEXP-11b(7) and CFEXP-11b(6), respectively.

FIG. 35 shows the X-ray diffraction spectrum for the ferritic (matrix) phase of the CFEXP-11b alloy.

FIGS. 36A and 36B shows backscatter-mode scanning electron micrographs (SEMs) of the microstructure of CFEXP-11 alloys.

FIG. 37 shows a backscatter-mode scanning electron micrograph (SEM) of the microstructure of a CFEXP-11 alloy with additional hard precipitates.

FIG. 38 is a plot of the ASTM G65 results for various exemplary alloys of this disclosure.

The figures are not intended to be exhaustive or to limit the invention to the precise form disclosed. It should be understood that the invention can be practiced with modification and alteration, and that the invention be limited only by the claims and the equivalents thereof.

DETAILED DESCRIPTION OF THE EMBODIMENTS OF THE INVENTION

Some embodiments are described herein in terms of structural sites. In these embodiments some components occupy solvent sites and others occupy primary solute sites. In further alloys, further components occupy secondary solute sites and in some cases components occupy tertiary solute sites. In many embodiments, the primary solute elements are defined as the solute which are larger than the solvent elements. For example, the primary solute elements may be approximately as at least 5% larger than the solvent elements. FIG. 1A is a table illustrating atomic radii of various elements that may serve as components in various alloys according to some embodiments of the invention.

In some embodiments of the invention, a class or group of compositions is determined using two criteria. In these embodiments, the first criteria is that the primary solute elements are larger than the solvent element, and the second criteria is that the thermodynamic properties of the compositions vary from those that would be predicted from the constituent elements alone. As an example of the first criteria, the primary solute element may comprise an element that is at least approximately 10% larger than the solvent element.

In one embodiment, a first class of alloys that satisfy these criteria may be formed when the solvent elements comprise transition metals ranging in atomic sizes from approximately 1.27 to 1.34 Å. As illustrated in FIG. 1A, some of these candidate elements may comprise V, Cr, Mn, Fe, Co, Ni, or Cu, for example. In this embodiment, some bulk metallic glasses may be formed by the addition of a larger primary solute element having an atomic size at least approximately 10% larger than the size of the solvent element. In this embodiment, these primary solute elements range from elements having atomic radii of at least about 1.41 Å for solvent elements having atomic radii of approximately 1.27 Å to elements having atomic radii of at least about 1.47 Å for solvent elements having atomic radii of 1.34 Å. For example, for Cu as a solvent, some possible candidate primary solutes comprise Mo, Pd, W, Ag, Al, Ti, or larger elements. Compositions formed according to this embodiment may further accommodate secondary or tertiary solute elements comprising metalloids or nonmetal elements. For example, such elements might comprise C, B, Si, P, N, or S. In further embodiments, this range of compositions may be more precisely defined according to certain thermodynamic properties.

In these embodiments, the second criteria for the class of compositions is satisfied when the alloys have a low liquid energetic state in comparison with the energy of the solid-state. For example, deep eutectics may be used as an experimental measure of the thermodynamic strength of the liquid in relation to the potential solid phases which it can form. In some embodiments, these energy comparisons may be performed by quantifying the eutectics of the compositions using a comparison between the actual melting or liquidus temperature of a specific alloy is compared to a calculated predicted liquidus temperature of the alloy. In these embodiments, the calculated liquidus temperature may be determined using a rule of mixtures type equation using the atomic percentages of the component elements and their respective pure melting temperature. For example, the calculated liquidus temperature T_(c) is determined according to the equation T_(c)=Σx_(i)T_(i) where x_(i) is the at. % of the component i and T_(i) is its pure melting temperature. For example, alloys within the compositional ranges of some embodiments of the invention may have calculated liquidus temperatures, T_(c), that are at least approximately 5% greater than the actual melting temperatures of the alloys. In further embodiments, different ratios between actual and calculated melting temperatures may be used. For example, as described herein some embodiments may comprise alloys having some degree of crystallinity, for example some alloys may comprise a micro or nanocrystalline alloys. Alloys within these embodiments may have calculated temperatures that are, for example, at least approximately 2% or 3% greater than the actual melting temperatures of the alloys. In still further embodiments, even deeper eutectics might be desirable for some applications, such as situations where molten alloys will experience lower than typical cooling rates. Alloys within these embodiments may have calculated temperatures that are, for example, at least approximately 7% or 8% greater than the actual melting temperatures of the alloys.

In some embodiments, the components of alloys may occupy distinct topological sites within the alloy. For example, a larger primary solute element may act as a centralized cluster site for solvent atoms to bind to during cooling. In these embodiments, these clusters allow the formation of a non-translational atomic packing scheme which resists crystallization. Furthermore, these larger solute atoms may generate elastic strain energy in an emerging crystalline embryo lattice composed of solvent elements and increase the likelihood for such an embryo to re-dissolve instead of acting as a seed for crystallization. In some instances, the topologies of these embodiments further allow secondary and tertiary solute elements to occupy interstitial sites that occur between the dense packing clusters. In some cases, these secondary or tertiary solute elements may create strong chemical interactions with the solvent elements.

In one embodiment, a class of metallic glass forming alloys comprises transition metal solvents with atomic radius sizes ranging from 1.27 to 1.34 Å. In this embodiment, primary solute sites may make up between 3 to 20 at. % of the alloy composition. These primary solute sites may be occupied by elements with atomic radii that are at least approximately 10% larger than those of the solvent. This embodiment may further comprise secondary solute sites that comprise approximately 10 to 25 at. % of the alloy composition. These secondary solute sites may be occupied by metalloid or nonmetal elements, for example C, B, Si, P, N, or S. The alloys within this embodiment further comprise alloys having melting temperatures that are at least approximately 5% less than a theoretical melting temperature calculated using a sum of the pure melting temperature of the components of the alloy weighted by their atomic percentages. FIGS. 1B through 1I illustrates some characteristics of examples of such alloys. In these figures the alpha parameter is determined according to the formula

${\alpha = \frac{\sum\; {x_{i}T_{i}}}{T_{l}}},$

where x_(i) is atomic percent of the ith element, T_(i) is the melting temperature of ith element, and T_(l) is the liquidus temperature of the alloy. As these figures illustrate, alloys that form amorphous structures tend to occur in ranges described herein.

In some alloys within this class, the number of available—or occupied—solute sites may vary according to various characteristics of the components. For example, the available secondary solute site may be somewhat dependent on characteristics of the primary solute or the solvent. For example, a primary solute that has a radius approximately 15% larger than that of the solvent may allow different secondary solutes or different amounts of secondary solutes to be used while still retaining metallic glass forming characteristics.

In a further embodiment of the invention, a second class of alloys may comprise alloys having solvent elements with atomic sizes in the range of 1.39 to 1.58 Å. For example, solvent elements within this second class may comprise Al, Ti, Zr, Nb, or Mo. In some instances, alloys within this class can accommodate a tertiary solute element in addition to primary and secondary solute elements. In this embodiment, primary solute sites may make up approximately 10 to 30 at. % of the alloy composition. These primary solute sites may be occupied by metallic elements having atomic radii that are at least approximately 5% smaller than the solvent elements. These alloys may further comprise elements making up 2 to 10 at. % of the alloy composition and occupying secondary solute sites. In some embodiments, these secondary solute elements may comprise elements having atomic radii that are at least approximately 5% larger than the solvent elements. In further embodiments, these alloys may further comprise elements making up 5-20 at. % of the alloy composition and occupying tertiary solute sites. These elements occupying tertiary solute sites may comprise metalloid or nonmetal elements such as C, B, Si, P, N, or S. Similarly to the first class of alloys, the alloys of these embodiments may be further defined according to their melting temperatures, wherein their melting temperature is below a predetermined percentage of a theoretical integer calculated using a weighted sum of the pure melting temperatures of the alloy's components. For example, in some embodiments the alloys may be defined according to a melting temperature that is at least approximately 5% less than such a theoretical temperature. In some embodiments, the addition of this tertiary solute element may increase packing density and thereby further increase viscosity of the alloy.

In further embodiments of the invention, the described alloys may be modified to produce alloys forming micro or nanocrystalline structures. For example, the relative sizes or amounts of the solvents or solutes may be varied to promote such formations. For example, the use of 1-2% more of a solvent may result in an alloys that forms a nanocrystalline or fine-grained structure instead of an amorphous structure. Additionally, the temperature requirements of some embodiments may be relaxed so that alloys having slightly higher melting temperatures, such as 2% less than the theoretical melting temperature, may be investigated for micro or nanocrystalline properties. In still further embodiments, bulk metallic glass alloys may be used to form micro, nanocrystalline or partially crystalline alloys without modification. For example, alloys within the above classes may be cooled at different rates or under different conditions to allow at least some crystallinity in the alloy.

FIGS. 2 through 5 are x-ray diffraction spectrograms of alloys determined according to an embodiment of the invention. As discussed herein, in some applications may be desirable to provide compositions that are partially amorphous and partially nanocrystalline. For example, these coatings may be useful in wear and corrosion resistant twin wire arc spray coatings. In some applications, the coating may benefit from having some limited amount of crystallinity in the coating to act as a binder phase for the remaining hard amorphous particles.

FIG. 2 is an x-ray diffraction spectrogram illustrating a twin wire arc spray coating having the following composition:

Element Fe Cr Mo C B W Ni wt percent 62 13 12 2.2 2.2 3.8 4.8 (atomic (56.3) (12.7) (6.3) (9.3) (10.3) (1) (4.1) percent)

In the illustrated coating, an amorphous phase fraction of approximately 75-85% was formed in the composition. In this composition, the Fe, Cr, and Ni occupy solvent sites, the Mo and W occupy primary solute sites, and the C and B occupy secondary solute sites. Accordingly, in the illustrated embodiment, elements occupying solvent sites comprise approximately 73 at. % of the alloy; elements occupying primary solute sites comprise approximately 7.3 at. % of the alloy; and elements occupying secondary solute sites comprise approximately 19.6 at. % of the alloy. In further embodiments, the specific elements occupying the topological sites may vary without significantly changing the atomic percentages of elements occupying those top logical sites. For example, in a further embodiment, an alloy may be formed by reducing the percentage of chromium while increasing the percentage of nickel to form an alloy having a melting temperature that is approximately 5% less than the calculated rule-of-mixtures melting temperature. In still further embodiments, the percentage of occupied sites may vary. For example, the atomic percentages of elements occupying the secondary solute sites may be increased at the expense of the elements occupying the solvent sites to form an alloy having a melting temperature that is approximately 3% less than the calculated rule-of-mixtures melting temperature.

FIG. 3 is an x-ray diffraction spectrogram illustrating a twin wire arc spray coating having the following composition:

Element Fe Cr Nb B Ni Si Mn wt 65.6 14.5 8.6 4.2 4.8 1.1 1.2 percent (atomic (56.5) (13.4) (4.5) (18.7) (3.9) (1.9) (1.1) percent) The illustrated composition has an amorphous phase fraction of approximately 45-55%. In this composition, the Fe, Cr, Ni, and Mn occupy solvent sites, the Nb occupies primary solute sites, and the Si and B occupy secondary solute sites. Accordingly, in the illustrated embodiment, the elements occupying the solvent sites make up approximately 74.9 at. % of the composition; elements occupying the primary solute sites make up approximately 4.5 at. % of the composition; and elements occupying secondary solute sites comprise approximately 20.6 at. % of the composition. As described herein, some variations of this alloy might comprise substituting similarly sized elements at appropriate topological sites, such as a substituting Ga for Ni; other variations of this alloy might comprise increasing or decreasing the atomic percentages of the various sites, such as decreasing or increasing the atomic percent of primary solute site elements by 1-5% and increasing or decreasing the atomic percent of secondary solute site elements by a corresponding amount.

FIG. 4 is an x-ray diffraction spectrogram illustrating a twin wire arc spray coating having the following composition:

Element Fe Cr Nb B Si Mn wt percent 65.9 24.6 4.6 2.2 1.5 1.2 (atomic percent) (59) (23.9) (3) (10.3) (2.7) (1.1) The illustrated composition has an amorphous phase fraction of approximately 35-45%. In this composition, the Fe, Cr, and Mn occupy solvent sites, the Nb occupies primary solute sites, and the Si and B occupy secondary solute sites. Accordingly, in the illustrated embodiment, the elements occupying the solvent sites make up approximately 84 at. % of the composition; elements occupying the primary solute sites make up approximately 3 at. % of the composition; and elements occupying secondary solute sites comprise approximately 14 at. % of the composition.

FIG. 5 is an x-ray diffraction spectrogram illustrating a twin wire arc spray coating having the following composition:

Element Fe Cr C B W Nb wt percent 67.3 9.6 2.1 1.6 8.8 10.6 (atomic percent) (64.3) (9.8) (9.3) (7.9) (2.6) (6.1) In this composition, the Fe and Cr occupy solvent sites, the Nb and W occupy primary solute sites, and the C and B occupy secondary solute sites. The illustrated composition has an amorphous phase fraction of approximately 0-20%.

In general, amorphous phase fraction and coating hardness will vary according to varying spray parameters. In the embodiments illustrated in FIGS. 2-5, the coating hardness as range from approximately between 800 and 1100 Vickers hardness. The particle hardness as our functions of the material compositions and not the coating porosity or inter particle adhesion. Typical embodiments of amorphous or nanocrystalline alloys formed within these classes have hardnesses that exceed 1200 Vickers.

FIGS. 6 and 7 are figures comparing known materials to the performance of an alloy according to an embodiment of the invention. In these figures, Fe_(67.5)Cr_(9.6)C_(2.1)B_(1.6)W_(8.8)Nb_(10.6) was compared to a tungsten carbide/cobalt (WC/CO) having 88% at. % WC and 12 at. % Co; a first Fe-based fine grain coating comprising Fe_(balance)C_(.04-.06)Si_(.6-1.5)Cr₂₅₋₃₀Ni₅₋₇Mn_(1.2-2.4)B_(3.2-3.7) (Alloy 1); and a second Fe-based fine grain coating comprising Fe_(balance)Cr_(<25)Mo_(<15)B_(<5)W_(<5)C_(<2)Mn_(<2)Si_(<2) (Alloy 2). In these comparisons, Fe_(67.5)Cr_(9.6)C_(2.1)B_(1.6)W_(8.8)Nb_(10.6) and the two other Fe-based alloys were deposited on a surface as under a twin wire arc spray coating. Due to the properties of WC/Co, this material was deposited using a high velocity oxygen fuel thermal spray process. As these results demonstrate, embodiments of this invention may serve as superior materials for a variety of applications requiring hardness and wear resistance. For example, some embodiments of this invention may serve as superior materials for bearing coatings, or for bearings themselves.

FIG. 6 demonstrates the results of a volume loss comparison using the ASTM G77 metal sliding wear test. As the figure demonstrates, Fe_(67.5)Cr_(9.6)C_(2.1)B_(1.6)W_(8.8)Nb_(10.6) had about a 0.07 mm³ volume loss in the test, while WC/Co had about a 0.13 mm³ volume loss and Alloy 1 and 2 each demonstrated about a 0.17 mm³ volume loss. As these results demonstrate, Fe_(67.5)Cr_(9.6)C_(2.1)B_(1.6)W_(8.8)Nb_(10.6) demonstrated about an 86% improvement over WC/Co and about an 142% improvement over Alloys 1 and 2. As described herein, similarity in structures between this embodiment and other embodiments of the invention are expected to result in similar improvements.

FIG. 7 demonstrates the results of a coefficient of friction comparison using the ASTM G77 metal sliding wear test. As the figure demonstrates, Fe_(67.5)Cr_(9.6)C_(2.1)B_(1.6)W_(8.8)Nb_(10.6) has a coefficient of friction of about 0.53, while WC/Co and Alloy 1 each have a coefficient of friction of about 0.61, and Alloy 2 has a coefficient of friction of about 0.65. As these results demonstrate, Fe_(67.5)Cr_(9.6)C_(2.1)B_(1.6)W_(8.8)Nb_(10.6) demonstrated about a 15% improvement over WC/Co and Alloy 1, and a 23% improvement over Alloy 2. As described herein, similarity in structures and properties between this embodiment and other embodiments of the invention are expected to result in similar improvements.

FIG. 8 shows the results of a galvanic potential comparison between an embodiment of the invention and a comparison alloy. In this test, Fe_(65.9)Cr_(24.6)Nb_(4.6)B_(2.2)Si_(1.5)Mn_(1.2) was compared to Fe_(balance)C_(.04-.06)Si_(.6-1.5)Cr₂₅₋₃₀Ni₅₋₇Mn_(1.2-2.4)B_(3.2-3.7) in a seawater galvanic cell with 316 stainless steel serving as a reference electrode. The alloy according to an embodiment of the invention demonstrated a galvanic potential of about −275 mV as compared to about −375 mV for Fe_(balance)C_(.04-.06)Si_(.6-1.5)Cr₂₅₋₃₀Ni₅₋₇Mn_(1.2-2.4)B_(3.2-3.7). These results demonstrate the superiority of some embodiments of the invention in corrosive environments, such as seawater. The results demonstrate that some embodiments of the invention have potentials similar to that of 400 series stainless steels. Accordingly, embodiments of the invention may serve as superior wear resistant coatings in applications such as ship hulls where traditional Fe-based coatings, even corrosive resistant coatings such as Fe_(balance)C_(.04-.06)Si_(.6-1.5)Cr₂₅₋₃₀Ni₅₋₇Mn_(1.2-2.4)B_(3.2-3.7), degrade too rapidly.

In various embodiments, many different materials may be formed using the methods described herein. For example, bulk metallic glass forming materials may be determined according to the formula Fe₆₂₋₆₆Cr₁₃₋₂₅(Mo,Nb)₄₋₁₂(C,B)_(2.2-4.4)Ni_(0-4.8)Si_(0-1.5)Mn_(0-1.2)W_(0-3.8), and particularly according to the formulae Fe₆₂₋₆₆Cr₁₄₋₁₆Nb₈₋₁₀B_(4-4.4)Ni_(3-4.8)Si_(0-1.1)Mn_(0-1.2) and Fe₆₀₋₆₆Cr₂₀₋₂₅Nb₄₋₅B₁₋₃Si_(1-1.5)Mn₁₋₂. In further embodiments, composite materials may be formed by combining components that are formed according to these formulae.

As described herein, adjusting some parameters may result in materials that form nanocrystalline or fine grained structures. For example, such nanocrystalline or fine grained structure may comprise materials defined by the formula Fe₆₇₋₆₉Cr_(9.6-10.9)(Mo,Nb)_(9.2-10.6)C_(1.4-2.1)B_(1.6-1.8)Si_(0-0.2)Ti_(0-0.2)W_(7.3-9), and more particularly according to the formulae Fe₆₇₋₆₉Cr_(9.6-10.9)C_(1.4-2.1)B_(1.6-1.8)W_(7.3-9)Nb_(9.2-10.6) and Fe₆₇₋₆₉Cr_(9.6-10.9)Mo_(4-5.3)C_(1-4-2.1)B_(1.6-1.8)W_(7.3-9)Nb_(4-5.3). In further embodiments, composite materials may be formed by combining components that are formed according to these formulae. In still further embodiments, other amorphous forming materials may be similarly modified to result in materials that form nanocrystalline or fine grained structures.

In additional embodiments, composite materials may be made that tend to form partially amorphous and partially nanocrystalline or fine grained structures. For example, one or more components defined by the above formulae for amorphous structured materials may be combined with one or more components defined by the above formulae for nanocrystalline or fine grained structured materials. In a specific embodiment, such a material may comprise a mixture of components selected from the group comprising:

-   -   (1) Fe₆₂Cr₁₃Mo₁₂C_(2.2)B_(2.2)W_(3.8)Ni_(4.8),     -   (2) Fe_(65.9)Cr_(24.6)Nb_(4.6)B_(2.2)Si_(1.5)Mn_(1.2),     -   (3) Fe_(65.6)Cr_(14.5)Nb_(8.6)B_(4.2)Ni_(4.8)Si_(1.1)Mn_(1.2),     -   (4) Fe_(67.5)Cr_(9.6)C_(2.1)B_(1.6)W_(8.8)Nb_(10.6), and     -   (5) Fe_(63.4)Cr_(9.4)Mo_(12.5)C_(2.5)B_(1.8)W_(10.4).

As described herein, some alloys that have a tendency to form amorphous or partially amorphous structures in some conditions are likely to form fine-grained weld overlays. Accordingly, some embodiments of the invention demonstrate improved hardness and toughness in hardface welding applications. FIG. 9 is a scanning election microscope (SEM) image of an alloy according to an embodiment of the invention, Fe_(67.5)Cr_(9.6)C_(2.1)B_(1.6)W_(8.8)Nb_(10.6), demonstrating this fine grain structure in a weld overlay coating. FIG. 10 illustrates the results of a test comparing the alloy of FIG. 9 to a first Fe-based fine grain coating comprising Fe_(balance)C_(.04-.06)Si_(.6-15)Cr₂₅₋₃₀Ni₅₋₇Mn_(1.2-2.4)B_(3.2-3.7) (Alloy 1) and a second Fe-based fine grain coating comprising Fe_(balance)Cr_(<25)Mo_(<15)B_(<5)W_(<5)C_(<2)Mn_(<2)Si_(<2) (Alloy 2). As illustrated, the alloy according the embodiment of the invention demonstrates a mass loss of about 0.07 G, compared to about 0.14 G for Alloy 1 and about 0.26 G for Alloy 2. Accordingly, the alloy of the embodiment of the invention demonstrates around a 100% to 200% improvement over Alloys 1 and 2.

In some hardfacing applications, WC or other hard particles are used as reinforcing the weld overlay. For example, coarse hard carbide particles may be introduced into the weld bead as it is being deposited. Some embodiments of the invention allow enable hardfacing weld overlays to be formed using WC or other hard particle reinforcement without significant cracking or decreased toughness. Furthermore, when these embodiments are used for the matrix of such reinforced weld overlays, they retain the hardness and wear resistance described herein. FIG. 11 is an SEM image demonstrating the results of 1000 kg load Vickers indentation on a hardfacing weld overlay comprising a matrix of an alloy formed according to an embodiment of the invention and coarse carbide particles. In this test, Fe_(75.1)Cr₁₀Nb₁₀B_(4.65)Ti_(.25) was used as a matrix for coarse carbide particles where the coarse carbide particles constituted 50% by volume of the weld overlay. These test results demonstrate the toughness of some embodiments of the invention; even under a 1000 kg load Vickers indentation, there was no cracking at the interface between the carbide particles and the matrix. FIG. 12 is an SEM showing a portion of this interface. As this figure illustrates, the hard carbide particles reprecipitate at the interface as opposed to dissolving into the matrix, which would otherwise introduce brittleness into the matrix. FIG. 13 is a further illustration of the toughness of a carbide reinforced weld overlay according to an embodiment of the invention. FIG. 13A demonstrates the fine grain structure of a carbide reinforced weld overlay comprising Fe_(75.1)Cr₁₀Nb₁₀B_(4.65)Ti_(.25). FIG. 13B illustrates a further 1000 kg load Vickers indentation test, again demonstrating an absence of cracking at the interface between the carbide particles and the matrix.

Further embodiments of the invention comprise ranges of alloys that demonstrate precipitation of a substantial fraction of hard carbide particles in carbide reinforced weld overlays. In one of the embodiments, a range of alloys is defined by the formula: Fe₆₇₋₇₁Cr_(9.6-9.7)(Mo,Nb)_(8.8-10.6)C_(1.8-2.2)B_(1.4-1.6)W_(7.4-8.8). For example, the alloy discussed with respect to FIGS. 9 and 10 is an alloy within this embodiment. In a further embodiment, the range of alloys comprises alloys defined by the formula Fe₆₇₋₇₁Cr_(9.6-9.7)Mo_(8.8-10.5)C_(1.8-2.2)B_(1.4-1.6)W_(7.4-8.8). In further embodiments, an alloy may be made up of a plurality of components, wherein one or more of the components comprises alloys defined by these formulae. Materials formed according to these embodiments have typical hardnesses of 1300-1450 Vickers hardness throughout the entire microstructures.

In another embodiment of the invention, a material that is suitable for hard particle reinforcement weld overlays comprises a component defined by the formula Fe₄₃₋₅₄Cr_(5.7-7.2)(Mo,Nb)_(6.6-15.5)C_(1-1.3)B_(1-1.8)W_(9.98-28)Ti₁₋₇. In further embodiments, such a component may be defined by the formula Fe_(50.5-53.2)Cr_(6-7.2)Mo_(6.6-7.9)C_(1.3-1.6)B_(1-1.2)W_(25-26.6)Ti₃₋₅. In additional embodiments, a component of a material may be defined partially by the first formula and partially by the second. For example, a component might comprise Fe₅₂Cr_(5.7)Mo_(8.9)C_(1.1)W_(26.2)Ti_(6.1). In still further embodiments, an alloy comprises a plurality of components, wherein the components are each defined by one of the above formulae. Embodiments of the invention formed according to these formulae may demonstrate substantial precipitation of hard particles in reinforced weld overlay applications. For example, FIG. 14 is a SEM demonstrating the precipitation of WC particles in a slow quenched ingot having a matrix comprising Fe_(43.2)Cr_(5.7)Mo_(15.5)C_(1.8)B_(1.3)W_(27.5)Ti₅. FIG. 14 further demonstrates that alloys formed according to these embodiments retain a fine-grained microstructure even under slow cooling conditions. Materials formed according to these embodiments have typical hardnesses of 1300-1450 Vickers hardness throughout the entire microstructures.

In one embodiment of the invention, a material that demonstrates hard particle precipitation comprises a component defined by the formula Fe₅₄₋₇₅Cr_(9-14.4)Ni_(0-4.8)(Mo,Nb)_(7.9-19.7)C_(1-6-2.1)B_(13-4.6)W_(0-9.98)Ti_(0.25-7)Si_(0-1.1)Mn_(0-1.1). FIG. 15 demonstrates that a component comprising Fe_(54.6)Cr_(7.2)Mo_(19.7)C_(2.1)B_(1.1)W_(9.5)Ti₅ demonstrates precipitation of a high fraction of embedded hard particles during slow cooling. FIG. 15 further demonstrates the fine-grained nature of these embodiments that occur in non-amorphous phase forming conditions. In a further embodiment of the invention, materials may be formed having a component that is defined by the formula Fe₇₀₋₇₅Cr₉₋₁₀Nb₇₋₁₀B_(4-4.6)Ti_(.25-7), Fe₅₄₋₆₃Cr_(7.2-9.6)Mo_(8.6-19.7)C_(1-6-2.1)B_(1.1-1.7)W_(8.5-9.5)Ti₃₋₇. Additionally, in some embodiments, materials may be formed having components that comprise combinations of these formulae. Materials formed according to these embodiments have typical hardnesses of 1300-1450 Vickers hardness throughout the entire microstructures.

In further embodiments of the invention, materials may be formed that comprise mixtures of alloys formed according to the formulae described herein. For example, a material may be formed comprising a plurality of components that are defined by the formulae Fe₅₄₋₇₅Cr_(9-14.4)Ni_(0-4.8)(Mo,Nb)_(7.9-19.7)C_(1-6-2.1)B_(1.3-4.6)W_(0-9.98)Ti_(0.25-7)Si₀₋₁₁Mn_(0-1.1) and Fe₄₃₋₅₄Cr_(5.7-7.2)(Mo,Nb)_(6.6-15.5)C_(1-1.3)B_(1-1.8)W_(9.98-28)Ti₁₋₇. In a specific embodiment, a material comprises a mixture of one or more of the following components:

-   -   (1) Fe_(67.5)Cr_(9.6)Mo_(5.3)C_(2.1)B_(1.6)W_(8.8)Nb_(5.3),     -   (2) Fe₆₉Cr_(10.9)Nb_(9.2)B_(1.8)C₁₋₄W_(7.3)Si_(0.2)Ti_(0.2),     -   (3) Fe_(67.5)Cr_(9.6)Mo_(10.5)C_(2.2)B_(1.6)W_(8.8),     -   (4) Fe_(70.9)Cr_(9.7)Mo_(8.8)C_(1.8)B_(1.4)W_(7.4),     -   (5) Fe_(43.2)Cr_(5.7)Mo_(15.5)C_(1.8)B_(1.3)W_(27.5)Ti₅,     -   (6) Fe_(50.5)Cr_(7.2)Mo_(7.9)C_(1.6)B_(1.2)W_(26.6)Ti₅,     -   (7) Fe_(53.2)Cr_(7.3)Mo_(6.6)C_(1.3)B₁W_(25.6)Ti₅,     -   (8) Fe_(50.3)Cr_(7.2)Nb_(7.9)C_(2.6)B_(1.2)W_(25.8)Ti₅,     -   (9) Fe_(57.2)Cr_(7.3)Mo_(6.6)C_(1.3)B₁W_(25.6)Ti₁,     -   (10) Fe_(51.2)Cr_(7.3)Mo_(6.6)C_(1.3)B₁W_(25.6)Ti₇,     -   (11) Fe_(54.6)Cr_(7.2)Mo_(19.7)C_(2.1)B_(1.1)W_(9.5)Ti₅,     -   (12) Fe_(67.4)Cr_(9.6)Mo_(9.4)C_(1.8)B₂W_(8.8)Ti₁,     -   (13) Fe₆₃Cr_(9.6)Mo_(8.6)C_(1.6)B_(1.7)W_(8.5)Ti₇,     -   (14) Fe_(70.2)Cr_(9.6)Mo_(8.7)C_(1.7)B_(1.4)W_(7.4)Ti₁,     -   (15) Fe₆₆Cr₉Mo_(8.2)C_(1.6)B_(1.3)W_(6.9)Ti₇,     -   (16) Fe_(75.1)Cr₁₀Nb₁₀B_(4.65)Ti_(0.25),     -   (17) Fe_(74.6)Cr_(9.9)Nb_(9.9)B_(4.6)Ti₁,     -   (18) Fe₇₀Cr_(9.3)Nb_(9.3)B_(4.4)Ti₇,     -   (19) Fe_(64.9)Cr_(14.4)Nb_(8.5)B_(4.8)         Ni_(4.1)Ti₁Si_(1.1)Mn_(1.2),     -   (20) Fe₆₁Cr_(13.5)Nb_(7.9)B_(4.5)     -   (21) Fe_(63.8)Cr_(9.6)Nb_(11.7)C_(2.1)B_(1.8)W₁₀Ti₁,     -   (22) Fe_(62.3)Cr_(9.6)Nb_(9.6)C_(1.9)B_(1.5)W_(8.1)Ti₇.

In a process according to one embodiment of the invention, coarse hard particles are combined with a hard matrix material comprising components described herein. This process comprises melting a component as described herein over a layer of coarse particles. For example, an arc melter may be used to melt a matrix material over a bed of coarse WC particles. In some embodiments, although melted WC may have a tendency to reprecipitate, it is desirable to minimize the amount of WC that dissolves into the melted matrix. In one embodiment, the coarse particles are disposed on a cooling body, such as a grooved hearth. For example, a water-cooled grooved copper hearth may be used. In this embodiment, the coarse particles are kept at a lower temperature to increase their resistance to dissolution. Accordingly, in these embodiments, the WC particles are allowed to metallurgically bind to the matrix without substantially dissolving into the matrix.

In particular experiments, this procedure was conducted using 30%, 40%, and 50% by weight coarse tungsten carbide particles, wherein the remaining weight percentages comprised a matrix material comprising components described herein. FIGS. 16 and 17 are SEM images demonstrating typical results of these experiments. FIG. 16 illustrates a typical result where 4-8 mesh 80-20 WC/Co was used as the hard particle, forming a composite material: Fe_(37.6)Cr₅Nb₅C_(L8)B_(2.4)W_(42.2)Co₆. As this figure indicates, the matrix forms a metallurgical bond with the WC/Co particle without substantially dissolving the particle into the matrix. FIG. 17 illustrates a typical result where 4-8 mesh 88-12 WC/Co particles served as the hard particle, forming a composite material: Fe_(52.7)Cr₇Nb₇C₁B_(3.3)W₂₃Co₆. This figure also demonstrates a metallurgical bond between the WC/Co particle and the matrix, without substantial dissolution of the particle into the matrix. The materials formed according to this embodiment are Fe and W based compositions comprising composite materials of WC hard particles embedded in a hard matrix. In these experiments, the Vickers hardness of the WC is approximately 1400, while the matrix demonstrated Vickers hardnesses of approximately 1200 due to some dissolution of the coarse particles into the matrix. The materials also demonstrate resistance to cracking at the interface between the particles and the matrix. Accordingly, these material are well-suited for applications where both extreme impact and extreme abrasive wear occur. In some embodiments, these materials may be pre-formed for use as components in other applications. As the materials cool, they may contract. Accordingly, the cooling surfaces, such as the grooved hearth, will typically be adjusted for such contractions.

In some embodiments, these composite materials may be formed using components defined by the formula (Fe_(54.6-75.3)Cr_(7.2-24.6)Mo_(0-19.7)C_(0-2.3)B_(1.5-4.7)W_(0-9.5)Nb₀₋₁₀Ti₀₋₇Si_(0-1.5)Mn_(0-1.2))×(W_(76.8-84.5)C_(3.2-3.5)Co₁₂₋₂₀)_(100-x) where x=50-70. In these embodiments, a matrix material may therefore be defined by the formula Fe_(54.6-75.3)Cr_(7.2-24.6)Mo_(0-19.7)C_(0-2.3)B_(1.5-4.7)W_(0-9.5)Nb₀₋₁₀Ti₀₋₇Si_(0-1.5)Mn_(0-1.2). In some specific embodiments, a composite material comprises one or more components defined by the formulae:

-   -   (1) Fe_(38.2)Cr₅Mo_(13.8)C_(2.7)B_(1.2)W₃₂Ti_(3.5)Co_(3.6)     -   (2) Fe_(27.2)Cr_(3.6)Mo_(9.9)C_(2.9)B_(0.9)W₄₇Ti_(2.5)CO₆     -   (3) Fe_(38.2)Cr₅Mo_(13.8)C_(2.7)B_(1.2)W₃₂Ti_(3.5)Co_(3.6)     -   (4) Fe₃₂Cr_(4.6)Mo₅C_(2.6)B_(0.8)W_(42.5)Ti_(2.5)Co₁₀     -   (5) Fe_(52.7)Cr₇Nb₇C₁B_(3.3)W₂₃CO₆     -   (6)         Fe_(46.2)Cr_(17.2)Nb_(3.2)C_(1.1)B_(1.5)W_(25.3)Ti_(3.2)Si_(1.1)Mn_(0.8)Co_(3.6)     -   (7)         Fe₄₉Cr_(6.5)Nb_(6.5)C_(1.1)B_(3.1)W_(25.3)Co₆Ti_(4.9)Co_(3.6)     -   (8) Fe_(37.6)Cr₅Nb₅C_(1.8)B_(2.4)W_(42.2)CO₆

In further embodiments, other materials disclosed herein may serve as suitable matrix materials. For example, the compounds described above with respect to weld overlay applications may serve as suitable matrix materials for these composite materials.

As described herein, a variety of elements may occupy solvent sites in various embodiments of the invention. For example, both Fe and Ni have an atomic radius of 128 Å. Accordingly, Ni may be substituted for some or all of an amount of Fe in the materials and components described herein. For example, in the material described with respect to FIG. 3, Fe_(65.6)Cr_(14.5)Nb_(8.6)B_(4.2)Ni_(4.8)Si_(1.1)Mn_(1.2), arbitrary amounts of Ni may be substituted for arbitrary amounts of Fe, such that the melting temperature of the resultant alloy remains at least approximately 5% less than the melting temperature predicted by a rule of mixtures. In some embodiments, these materials containing Ni may be particularly well-suited for brazing applications. In particular embodiments, these brazing alloys comprise alloys having components defined by the formula (Ni,Fe)₅₀₋₉₅(Si,B,P)₀₋₂₀Cr₀₋₃₅. In further embodiments the relationship between Ni and Fe may be further defined according to the methods and processes described herein, such as inspection of melting temperatures compared to rule of mixture melting temperatures. In a specific embodiment, such a braze material comprises at least one component selected from the group comprising Ni₅₂B₁₇Si₃Fe₂₈, Ni₅₅B₁₈Cr₄Fe₂₄, Ni₅₄B₁₄Si₄, Cr₄Fe₂₄, Ni₅₂B₂₀Fe₂₈, and Fe₄₃Cr₃₃Ni₁₀B₁₄.

In additional embodiments, the alloys may further contain additives to enhance or introduce various features. For example, small amounts of Al, Ca, Y, misch metal, or other materials may be added as oxygen getters. In the above formula, the addition of these oxygen getters results in the formula (Ni,Fe)₅₀₋₉₅(Si,B,P)₀₋₂₀Cr₀₋₃₅(Al, CA, Y, misch)₀₋₁, or more particularly (Ni,Fe)₅₀₋₉₅(Si,B,P)₀₋₂₀Cr₀₋₃₅(Al, CA, Y, misch)_(0-0.2).

In further embodiments, binder materials such as Al may be added to the compositions described herein. For example, the materials employed in twin wire arc spray methods described herein may be wrapped with a sheath such as mild steel, stainless steel, nickel, nickel chrome, or aluminum such that the resultant coating shows an increase in bond strength. In some embodiments, an amorphous or nanocrystalline coating produced using the twin wire arc spray method manufactured using a mild steel, stainless steel, nickel, or nickel chrome sheath resulted in bond strengths exceeding 8000 psi as measured by ASTM C 633. In further embodiments, wrapping an Al sheath around a solid or cored wire containing Ni-base materials described herein also may result in increased bond strengths. In additional embodiments, Al may be added to any material described herein in a range of concentrations. In these embodiments, the other elements of the material will typically be reduced by a proportional amount so maintain their relative concentrations. For example, Al may be added in concentrations of 0.5-10% to form materials having components defined by:

-   -   (1)         (Fe₆₂₋₆₆Cr₁₃₋₁₄(Mo,Nb)₈₋₁₂(C,B)_(4.2-4.4)Ni_(4.8)Si_(0-1.1)Mn_(0-1.2)W_(0-3.8))_(100-x)Al_(x)     -   (2)         (Fe₆₇₋₆₉Cr_(9.6-10.9)(Mo,Nb)_(9.2-10.6)C_(1-4-2.1)B_(1.6-1.8)Si_(0-0.2)Ti_(0-0.2)W_(7.3-9))_(100-x)Al_(x)     -   (3)         (Fe₆₇₋₇₁Cr_(9.6-9.7)Mo_(8.8-10.5)C_(1.8-2.2)B_(1.4-1.6)W_(7.4-8.8))_(100-x)Al_(x)     -   (4)         (Fe₄₃₋₅₃Cr_(5.7-7.2)(Mo,Nb)_(6.6-15.5)C_(1-1.3)B_(1.3-1.8)W_(9.98-28)Ti₁₋₇)_(100-x)Al_(x)     -   (5)         (Fe₆₁₋₇₅Cr_(9-14.4)Ni_(0-4.8)(Mo,Nb)_(7.9-11.7)C_(1-6-2.1)B_(1.3-4.6)W_(0-9.98)Ti_(0.25-7)Si_(0-1.1)Mn_(0-1.1))_(100-x)Al_(x)         where x ranges from 0.5% to 10%. In a specific embodiment,         increased bond strengths occur in some applications where         components are defined by the formula         Fe₆₅₋₆₇Cr₁₁₋₁₃Nb₄₋₆B₄₋₅Ni₄₋₆Si_(0-1.5)Mn_(0-1.5)Al₁₋₃. In         particular, the composition Fe₆₇Cr₁₃Nb₆B₄Ni₅Si₁Mn₁Al₂         demonstrated a bond strength exceeding 10,000 psi. Accordingly,         the addition of Al to materials described herein may further         increase the materials' utilities in applications requiring high         coating bond strength and abrasion resistance.

Certain materials disclosed in the present disclosure can be directed toward weld overlay materials. In some embodiments, although they are suitable for other weld overlay hardfacing applications, the materials serve as a superior weld overlay material for the protection of tool joints in oil and gas drilling operations.

Some embodiments comprise an iron-based alloy capable of forming a crack free hardbanding weld overlay coating on a curved substrate of 6″ or smaller without any pre-heating or slow cooling methods, resulting in a 60+ Rockwell C surface. In further embodiments, when welded, the alloy has a welded microstructure comprising a fine-grained ferritic matrix containing <10 μm Nb and W carbide precipitates. In still further embodiments, the alloys may be magnetic or non-magnetic in nature.

Particular embodiments comprise alloys falling within the range of alloys defined by the formula (In weight percent): Fe_(67.3-77.05)Cr₃₋₇Nb₄₋₇C_(0-5-1.4)B_(0.6-1.75)W_(9.5-15.45)Ti_(0-0.5)Si_(0-0.5)Mn₀₋₂Ni₀₋₂. Other embodiments comprise alloys falling within the range of alloys defined by the formula (In weight percent): Fe_(67.3-77.05)Cr₃₋₇Nb₄₋₇C_(0-5-1.4)B_(0.6-1.75)W_(9.5-15.45)Ti_(0-0.5)Si_(0-0.5)Mn₀₋₆Ni₀₋₃. A specific embodiment comprises the alloy given by the formula (In weight percent): Fe_(74.35)Cr₅Nb₄V₂B₁C_(0.8)W_(12.45) Si_(0.15)Ti_(0.25). Other embodiments comprise the alloy given by the formula (In weight percent): B_(1.15-1.25)C_(10-1.1)Cr_(4.8-5.0)Fe_(bal)Mn_(<1.0)Nb_(4.0-4.2)Si_(<1.0)Ti_(0.2-0.3)V_(1.95-2.05)W_(12.4-12.5). Other embodiments comprise the alloy given by the formula (In weight percent): B_(1.15-1.25)C_(1.0-1.1)Cr_(4.8-5.0)Fe_(bal)Mn_(<1.0)Nb_(.4.0-4.2)Si_(<1.0)Ti_(0.2-0.3)V_(0.40-0.60)W_(8.8-9.2).

FIG. 18 illustrates a metal inert gas (MIG) weld bead of an alloy implemented in accordance with an embodiment of the invention. Here, alloy 1800 comprised the alloy defined by the formula (In weight percent): Fe_(67.3-77.05)Cr₃₋₇Nb₄₋₇C_(0.5-1.4)B_(0.6-1.75)W_(9.5-15.45)Ti_(0-0.5)Si_(0-0.5)Mn₀₋₆Ni₀₋₃. The weld bead 1800 was applied to a 4140 steel 6″ diameter pipe 1801. As measured using a liquid dye penetrant, the weld bead shoed no cracking or cross-checking.

In one embodiment, a microstructure of an alloy by the formula (In weight percent): Fe_(74.35)Cr₅Nb₄V₂B₁C₀₋₈W_(12.45)Si_(0.15)Ti_(0.25) is provided. The microstructure of this alloy includes an optimized microstructure with a ferrite matrix having fine-grained niobium and tungsten based precipitates. These precipitates are less than about 10 μm on average and produce an alloy having a unique hardness and toughness. The matrix is a fine-grained ferritic/austentic matrix which is fully interconnected. The matrix is able to blunt cracking and provides toughness to the overall material The secondary phases and are extremely hard and are plentiful in the microstructure, forming up to 30% by volume fraction, but are isolated from each other by the interconnected matrix.

Three alloy compositions have been determined for manufacture into welding wires for hardbanding testing. The alloys have been determined from experimental results as part of an ongoing project to design hardbanding alloys, and subsequent laboratory analysis of potential alloys compositions. Initial laboratory results suggested these alloys as ideal candidates and the experimental welding trials have been conducted.

The alloy presented in this disclosure, namely, Fe_(74.35)Cr₅Nb₄V₂B₁C₀₋₈W_(12.45)Si_(0.15)Ti_(0.25), immediately showed promise as the alloy formed a crack free weld overlay on a 6″ round pipe without the use of a pre-heating step. Further analysis, including independent verification of a crack-free weld, and wear performance, indicated that the weld alloy represented a technological advance to currently used alloys and materials for use in oil and gas drilling.

The alloys presented in this disclosure offer many unique advantages to currently available weld overlay alloys, which when simultaneously utilized provide substantial benefit to the oil and gas drilling operation. Previously, no other single alloy could offer all these benefits to the hardbanding process and operation. Some of the advantages that embodiments of the invention present include the following.

First, crack-free as deposited welds: The alloys disclosed can be welded onto curved surfaces without the use of pre-heating or slow cooling techniques, and form a continuous crack free weld bead. The lack of pre-heating required is very advantageous not only because it eliminates an extra step in the process, but it prevents the possible deterioration of the inner polymer coating which is commonly used in drill pipes and is subject to failure when the pipe is pre-heated. Slow cooling is also a step which is generally unavailable to hardbanding done in the field, and it is advantageous if it is not required. Previously, these capabilities could be achieved only with weld overlay alloys that had substantially lower surface hardness levels.

Second, ability to be welded over itself and other weld beads without cracking: Weld overlays metallurgically bond to the substrate material and form a novel diluted alloy which is partially the original welding alloy and partially the substrate base material alloy. This dilution effect create different weld compositions depending upon the base metal that it is being welded onto. In the practice of oil drilling hardbanding it is common to re-weld over the top of a weld bead once it has partially worn away. In the case of many hardbanding alloys, this re-welding creates enough of a compositional shift in the weld when compared to welding atop of the original un-welded part, that cracking occurs in the re-weld whereas none occurred in the original weld. The alloys presented in this patent are have sufficient crack resistant such that they can be welded atop previous welds and experience no cracking. Previously, this capability could be achieved only with weld overlay alloys that result in substantially lower surface hardness levels.

Third, high hardness: The alloys described in this patent contain hardness levels of 60 Rockwell C or higher in the diluted condition when welded onto 4140 steel pipe under conditions similar to those used in the field application of hardbanding alloys for tool joints. Typical hardbanding alloys report 60+ Rockwell C values only when measured in the undiluted condition. However, in actual single pass weld overlays with significant dilution, which is the condition used for these applications, these alloys experience lower hardness values.

Fourth, improved wear resistance: The alloys described in this patent possess improved wear resistance compared to the previously most advanced hardbanding alloys used in oil and gas drilling operations. The wear resistance is measured using the ASTM G65 dry sand wear test. The wear loss of this alloy in the diluted condition (the condition typically used in the actual oil and gas drilling operations) was 0.1092 grams lost, significantly better than previous technologies which report un-diluted (condition resulting in lower wear losses, and not a condition used in the field) 0.12 g lost.

Fifth, the ability to absorb excess carbon with no or limited cracking: The alloys described in this patent are compositionally designed to form a high fraction of finely grained carbide precipitates. The thermodynamics inherent to these alloys allow for excess carbon to be absorbed into the weld without altering the advantageous microstructure, resulting in no or minimal cracking. This effect is advantageous in the hardbanding industry as a MIG carbide process is typically used to create hardbanding weld beads. In this process, WC/Co particles (˜1 mm in size) are fed into the weld bead as the weld is being made. This process creates a very difficult substrate to weld atop as there is a large concentration of W and C which will be introduced into the re-welded composition and microstructure. Previously used hardbanding alloys would experience drastic changes in microstructure and properties as a result of being re-welded onto this particular substrate. However, the designed chemistry of the alloy presented in this patent are flexible enough to absorb the excess carbon and tungsten and see relatively small changes in microstructure and properties. Thus, even when welded onto a un-worn MIG-carbide weld bead, they will experience only slight cross checking.

Sixth, optimal microstructure for limited casing wear: In drilling operations, the hardbanding weld beads constantly rub and wear against the outer casing. It is very critical that the hardbanding weld bead not wear away sufficiently against the casing so as to cause casing failure. Alloys which do not result in extreme casing wear are termed, ‘casing friendly’. Early hardbanding techniques such as MIG carbide, where coarse carbide grains were introduced into the weld, resulted in extreme casing wear and proved unacceptable in drilling operations where a casing was a requirement. The MIG carbide welds are formed of a soft steel matrix containing large carbide grains. The wear behavior is such that the steel quickly wears a way leaving the sharp carbide particles to gouge away at the casing. In the alloys presented in this patent, the carbide particles are very fine and evenly distributed so as not to cause highly localized regions of wear on the casing. Furthermore, the matrix is a hardened fine-grained structure, which exhibits hardening according to the Hall-Petch relationship. Thus, the casing will be in contact with a relatively smooth surface as opposed to a weld bead with sharp hard particles which locally wear and cause casing failure.

Some embodiments of hardbanding materials comprise alloys falling within the range of alloys defined by the formula (In weight percent): Fe_(65.3-79.95)Cr₃₋₇Ni₀₋₆Mn₀₋₆Nb_(3.5-7)V_(0-2.05)C_(0.5-1.5)B_(0.6-1.75)W_(7.5-15.45)Si_(0-1.0)Ti_(0-1.0)Al₀₋₄. Particular embodiments comprise alloy defined by the formulae (in weight percent): Fe_(65.3-79.95)Cr₅Ni₀₋₆ Mn₀₋₆Nb_(3.5-6)V₀₋₂C_(0.8-1.5)B_(0.8-1.4)W_(8.5-13.5)Si_(0.15)Ti_(0.25-1)Al₀₋₄; Fe_(bal)Cr_(4.8-5.2)Mn_(<1.1)Nb_(0.4.0-4.4)C_(1.0-1.1)V_(0.40-2.8)B_(0.8-1.25)W_(7.5-9.2)Si_(<1.0)Ti_(0.2-0.3); or Fe_(bal)Cr_(5.1)Mn_(1.1)Nb_(4.3)C_(1.1)V_(2.7)B_(0.8)W_(7.6)Si_(0.5)Ti_(0.2). Weight percents of various constituent elements in some exemplary embodiments falling within the range are listed in the following table 1:

TABLE 1 Exemplary alloy chemistries: Alloy ID Fe Cr Ni Mn Nb V C B W Si Ti Al H5A 71.35 5 0 2 4 2 0.8 1 13.45 0.15 0.25 0 H5B 67.3 5 0 6 4 2 0.85 1 13.45 0.15 0.25 0 H5C 71.3 5 2 0 4 2 0.85 1 13.45 0.15 0.25 0 H5D 67.3 5 6 0 4 2 0.85 1 13.45 0.15 0.25 0 H5E 65.3 5 2 6 4 2 0.85 1 13.45 0.15 0.25 0 H5F 65.3 5 6 2 4 2 0.85 1 13.45 0.15 0.25 0 H5G 72.65 5 0 0 4 2 1.3 1.2 13.45 0.15 0.25 0 H5H 72.65 5 0 0 4 2 1.5 1 13.45 0.15 0.25 0 H5I 72.85 5 0 0 4 2 1.5 0.8 13.45 0.15 0.25 0 H5J 72.15 5 0 0.5 4 2 1.1 1.4 13.45 0.15 0.25 0 H5K 77.3 5 0 0 4 2 0.8 1 9.5 0.15 0.25 0 H5L 75.5 5 0 0 4 2 1 1.1 11 0.15 0.25 0 H5M 73.25 5 2 0 4 2 0.85 1 11.5 0.15 0.25 0 H5N 75.25 5 0 0 6 2 0.85 1 9.5 0.15 0.25 0 H5O 75.25 5 2 0 4 2 0.85 1 9.5 0.15 0.25 0 H5P 75.3 5 2 0 4 2 1 0.8 9.5 0.15 0.25 0 H5Q 70.8 5 2 0.5 4 2 0.85 1 13.45 0.15 0.25 0 H5R 73.3 5 2 0 6 2 1 0.8 9.5 0.15 0.25 0 H5S 73.8 5 3 0.5 4 2 1 0.8 9.5 0.15 0.25 0 H5T 72.8 5 4 0.5 4 2 1 0.8 9.5 0.15 0.25 0 H5U 66.9 5 6 0 4 2 1.4 0.8 13.5 0.15 0.25 0 H5V 72.3 5 3 2 4 2 1 0.8 9.5 0.15 0.25 0 H5W 73.3 5 3 1 4 2 1 0.8 9.5 0.15 0.25 0 H5X 72.1 5 3 2 4 2 1.2 0.8 9.5 0.15 0.25 0 H5Y 71.9 5 3 2 4 2 1.4 0.8 9.5 0.15 0.25 0 H5& 70.1 5 3 2 4 2 1.2 0.8 11.5 0.15 0.25 0 H5Z 70.9 5 6 0 4 2 1.4 0.8 9.5 0.15 0.25 0 H7A 78.75 5 0 0 4 0.25 1 1.1 9.5 0.15 0.25 0 H7B 79 5 0 0 4 0 1 1.1 9.5 0.15 0.25 0 H7C 76.75 5 0 0 4 0.25 1 1.1 9.5 0.15 0.25 2 H7D 74.75 5 0 0 4 0.25 1 1.1 9.5 0.15 0.25 4 H7E 78.75 5 0 0 4 0 1 1.1 9.5 0.15 0.5 0 H7F 78.25 5 0 0 4 0 1 1.1 9.5 0.15 1 0 H7G 78.5 5 0 0 4 0.5 1 1.1 9.5 0.15 0.25 0 H7H 78.55 5 0 0 4 0 1.2 1.1 9.5 0.15 0.5 0 H7I 78.85 5 0 0 4 0.25 1.2 0.8 9.5 0.15 0.25 0 H7J 78.75 5 0 0 4 0 0.8 1.3 9.5 0.15 0.5 0 H7K 78.95 5 0 0 4 0.25 1 0.9 9.5 0.15 0.25 0 H7L 78.55 5 0 0 4 0.5 0.9 1.4 9 0.15 0.5 0 H7M 77.95 5 0 0 4 0.5 1 1.4 9.5 0.15 0.5 0 H7N 79.65 5 0 0 4 0 1.1 1.1 8.5 0.15 0.5 0 H7O 79.3 5 0 0 4 0 1 0.8 9.5 0.15 0.25 0 H7P 79.9 5 0 0 4 0 1 1.2 8.5 0.15 0.25 0 H7Q 79.95 5 0 0 4 0.25 1 0.9 8.5 0.15 0.25 0 H7R 79.75 5 0 0 4 0.25 1.1 1 8.5 0.15 0.25 0 H7S 79.85 5 0 0 3.5 0.25 1.1 0.9 9 0.15 0.25 0 H7T 78.65 5 0 0 4.5 0.25 1.1 1.1 9 0.15 0.25 0 H7U 78 5 0 0 4.5 0.5 1 1.1 9.5 0.15 0.25 0 H7V 78.75 5 0 0 4.5 0.25 1 1.1 9 0.15 0.25 0 H7W 79 5 0 0 3.5 0.5 1 1.1 9.5 0.15 0.25 0 H7X 78.75 5 0 0 4.5 0.25 1.1 1 9 0.15 0.25 0 H7Y 78.3 5 0 0 4.5 0.25 1.1 1.2 9 0.15 0.5 0 H7Z 78.25 5 0 0 4.5 0.25 0.9 1.2 9.5 0.15 0.25 0 CF-1 76.62 5.12 0 1.08 4.27 2.69 1.07 0.82 7.61 0.52 0.2 0

FIG. 19 is a diagram depicting an alloy design process 1900 according to certain aspects of the present disclosure. The alloy design process comprises a 4-component metallic glass modeling technique based on topology, liquidus temperature, chemical short range order and elastic strain to determine an amorphous forming epicenter composition. An amorphous forming composition epicenter 2010 and an associated amorphous forming composition range 2020 are shown in diagram 2000 of FIG. 20. Various aspects of such a 4-component metallic glass modeling technique are described above in the present disclosure and also in University of California, San Diego Ph.D dissertation “Modeling the Glass Forming Ability of Metals” by Justin Lee Cheney, which is incorporated by reference herein for all purposes. The modeling technique can be used to maximize the potential for amorphous forming ability for the design of an amorphous material 1920 having a metallic glass epicenter composition.

After determining an amorphous forming epicenter composition, a variant composition having a predetermined change in constituent elements from the amorphous forming epicenter composition is determined, and an alloy having the variant composition is formed and analyzed.

For example, a first or second variant technique 1930 or 1940 may be employed to design a thermal spray material (e.g., glass/crystal composite 1950) for use as a thermal spray wire or a fine-grained crystalline material (e.g., μm-structured crystalline 1960) for use as a weld overlay material, respectively.

A. Design of a Thermal Spray Material

The first variant technique 1930 for designing a thermal spray material (e.g., glass/crystal composite structures 1950) involves vitrification potential determination 1932 and solidification analysis 1934.

With regard to the vitrification potential determination 1932, in order to design glass/crystal composites, one or more variant compositions ranging from between about 5 and 10% atomic percent offset in constituent elements from an amorphous forming composition epicenter 2010 are chosen. As used herein, the term “about” means within normal manufacturing tolerances. This range is termed nanocrystalline/glass composite zone 2030 in diagram 2000 shown in FIG. 20. A variant composition in this nanocrystalling/glass composite zone can include one or more additional components that are not present in the amorphous forming epicenter composition. In certain embodiments, the variant composition includes between about 0.1 and 10% additional constituent that is not present in the amorphous forming epicenter composition.

The solidification analysis 1934 can be performed through a lab-based technique to simulate the cooling rate in thermal spray materials thus determined. In an exemplary setup 2108, an homogeneous alloy ingot is melted within an arc melter such as the one shown in FIG. 21 in a water cooled copper cavity 2107. When a fully molten copper plate 2105, termed the splat block, is dropped onto the liquid alloy ingot 2106, the liquid alloy ingot is rapidly cooled in the form of a thin sheet (between about 0.25 and 1 mm) in thickness. The resulting composite nanocrystalline/glass microstructure can be evaluated using any known structural analysis methods including, but not limited to, XRD and SEM analysis. Those variant compositions that satisfy certain conditions (e.g., hardness and structural integrity) are selected. Variant compositions designed and selected through the processes described above can be produced as thermal spray wires, for instance.

B. Design of a μm Crystalline Structure (Weld Overlay Material)

The second variant technique 1940 for designing a fine-grained crystalline material (e.g., μm-structured crystalline 1960) can involve a phase diagram prediction 1942 and a phase chemistry prediction 1944.

In the phase diagram prediction 1942, specific alloying elements are either added or subtracted to encourage an evolution of desired crystalline phases in the microstructure as illustrated by phase diagram 2200 shown in FIG. 22. The phase chemistry prediction 1944 can be used to model any shifts in elemental concentration of the liquid as primary crystallites nucleate.

Analysis of composition behavior is completed using specially designed experimental lab-based techniques to simulate the cooling rate of the weld. FIG. 23 illustrates an exemplary alloy formation and analysis procedure. In the procedure, an homogeneous alloy ingot is melted, e.g., within an arc melter in a water cooled copper cavity. Size of the homogenous alloy ingot being melted (“melt”) is preferably between about 10 and 20 g to ensure that the cooling rate closely matches that experienced in MIG welding. FIG. 24 is a diagram 2400 depicting liquid composition versus cooling curves for various constituent compositions. Certain variant compositions designed, analyzed and selected through the processes described above can be produced as welding wires, for instance.

FIGS. 25-38 illustrate the results of experiments performed on various additional embodiments of the invention. Exemplary alloy chemistries of these embodiments are listed in Table 2 below. Some of these alloys may have chemistries defined by the following formula: a balance of Fe; between 0-5.75 wt. % Cr; between 0-1.15 wt. % Mn; between 4-7 wt. % Nb; between 0-2.78 wt. % V; between 0.5-1.1 wt. % C; between 0.82-3 wt. % B; between 0-3.5 wt. % Mo; between 0-11.45 wt. % W; between 0-0.3 wt. % Ti; and between 0-5 wt. % Si. Additionally, some of these alloys may have chemistries defined by the following formula: a balance of Fe; between 0-5.75 wt. % Cr; between 0-1.15 wt. % Mn; between 4-7 wt. % Nb; between 0-2.78 wt. % V; between 0.5-1.1 wt. % C; between 0.82-3 wt. % B; between 0-3.5 wt. % Mo; between 0-11.45 wt. % W; between 0-0.3 wt. % Ti; and between 0-5 wt. % Si. In still further embodiments, a balance of Fe; between 0-6 wt. % Cr; between 0-6 wt. % Ni; between 0-2 wt. % Al; between 0-6 wt. % Mn; between 2-7 wt. % Nb; between 0-1 wt. % V; between 0.5-1.5 wt. % C; between 1.25-3 wt. % B; between 0-4 wt. % Mo or W; between 0-1 wt. % Ti; and between 0-1 wt. % Si. In yet further embodiments, the alloys may have chemistries defined by the following formula: a balance of Fe; between 4-6 wt. % Cr; between 0.8-1.2 wt. % Mn; between 4-5 wt. % Nb; between 0-1 wt. % V; between 0.6-1.1 wt. % C; between 1.25-2.25 wt. % B; between 2-4 wt. % Mo; between 0.1-0.5 wt. % Ti; and between 0.4-0.75 wt. % Si.

As described above, such alloy chemistries may be used in the production of welding wires for hardbanding applications or other welding applications. The chemistries may also be present in the final welds. The alloy compositions provided in Table 2 where created in the form of 10-20 g alloy ingots using a small bell jar (ABJ-338) arc melter. The specific compositions were produced by mixing together pure elemental granules, powders, and other feedstock and then melted completely in the arc melter under an argon atmosphere. To ensure complete mixing, the ingots were flipped and re-melted at least four times. No indication of incomplete melting was seen in any ingot microstructures.

TABLE 2 Exemplary alloy chemistries (in weight percent). Alloy # Fe Cr Nb Mo Ni V C B W Ti Si Mn CF-1 76.62 5.12 4.27 0 0 2.7 1.07 0.82 7.6 0.2 0.5 1.1 CF1-7 76.99 5.12 4.27 0 0 2.7 0.7 0.82 7.6 0.2 0.5 1.1 CF1-8 76.89 5.12 4.27 0 0 2.7 0.8 0.82 7.6 0.2 0.5 1.1 CF1-9 76.79 5.12 4.27 0 0 2.7 0.9 0.82 7.6 0.2 0.5 1.1 CFEXP-1 83.93 5 4.3 0 0 0.5 0.8 1.25 3 0.2 0.52 0.5 CFEXP-2 81.68 5 4.3 0 0 0.5 0.8 2.5 4 0.2 0.52 0.5 CFEXP-4 80.4 5 4.3 0 2 0.5 0.8 3 2 0.2 0.65 1.15 CFEXP-5 82.45 5 4.3 3 0 0.5 0.8 1.25 0 0.2 2 0.5 CFEXP-6 82.1 5 4 3.5 0 0.5 0.8 0.9 0 0.2 2 1 CFEXP-7 79.1 5 4 3.5 0 0.5 0.8 0.9 0 0.2 5 1 CFEXP-11a 82.95 5 4.3 3 0 0.5 0.8 1.75 0 0.3 0.4 1 CFEXP-11b 82.75 5 4.3 3 0 0.5 0.8 1.95 0 0.3 0.4 1 CFEXP-12 83.45 5 4.3 3 0 0.5 0.8 1.25 0 0.3 0.4 1 CFEXP-13 88 3 3 2 0 0.5 0.8 1 0 0.3 0.4 1 CFEXP-14 84 3 3 0 0 1.4 0.8 1.1 5 0.3 0.4 1 CFEXP-15 85.21 0 3.44 0 0 1.6 0.8 1.25 6 0.3 0.4 1 CrF-1 80.75 0 4 0 0 2 0.8 0.6 11.45 0.15 0.25 0 CrF-2 81.55 0 4 0 0 1 0.8 0.8 11.45 0.15 0.25 0 CrF-3 81.15 0 4 0 0 0 1 2 11.45 0.15 0.25 0 CrF-4 81.05 0 4 0 0 0 2 1.1 11.45 0.15 0.25 0 CrF-5 80.15 0 4 0 0 1 1 2 11.45 0.15 0.25 0 CrF-6 81.15 0 4 0 0 1 1 1 11.45 0.15 0.25 0 CrF-7 82.05 0 4 0 0 0 1.1 1 11.45 0.15 0.25 0

Alloy Group CF-1-CF1-9

As understood in the art, because of production variances, the final composition amounts of a welding wire or other material can differ from the exact desired chemistry. The alloys from Table 2 denoted CF-1, CF1-7, CF1-8, and CF1-9 represent four alloys produced with a similar chemistry as alloy CF-1 from Table 1, illustrating an example of possible ranges that may be obtained because of unavoidable production variation. Some embodiments may comprise compositions having the following elemental ranges: a balance of Fe; between 4-5.75 wt. % Cr; between 0.5-1.15 wt. % Mn; between 4-6 wt. % Nb; between 2-2.78 wt. % V; between 0.6-1.1 wt. % C; between 0.7-0.9 wt. % B; between 7-8 wt. % W; between 0.1-0.3 wt. % Ti; and between 0.25-0.75 wt. % Si. For example, the compositions may be welding wires, welds, or any metal alloy. Additionally, embodiments may comprise welding wires operable to create alloys having these ranges when used on various substrates.

Alloy Group CFEXP

Based on hardness measurements and microsctural analyses, several alloy chemistries (CFEXP-1, CFEXP-2, CFEXP-4, CFEXP-5, CFEXP-6, CFEXP-7, CFEXP-11, CFEXP-12, CFEXP-13, CFEXP-14, CFEXP-15) were manufactured in the form of 1/16″ cored welding wire. The CFEXP alloys were welded onto 4137 tool joints using welding parameters typical of the hardbanding process.

Some embodiments of invention comprise a composition of matter having the following compositional range: a balance of Fe; between 0-5 wt. % Cr; between 0-1.15 wt. % Mn; between 3-5 wt. % Nb; between 0.4-1.75 wt. % V; between 0.7-0.9 wt. % C; between 0.82-3 wt. % B; between 0-3.5 wt. % Mo; between 0-6 wt. % W; between 0.1-0.3 wt. % Ti; and between 0.25-5 wt. % Si. For example, such compositions may be welds, welding wires, or alloys. Additionally, some embodiments may comprise welding wires having compositions operable to produce welds having these alloy compositional ranges, or any other alloy composition disclosed herein

Several variations of the CFEXP-11 alloys were produced and are indicated in this disclosure as CFEXP-11a, CFEXP-11b (6), and CFEXP-11b (7). These alloy variations represent slight chemistry variations due to being produced in different manufacturing lots. The intended chemistry is CFEXP-11a. The difference between CFEXP-11b (6) and CFEXP-11b (7) are the arc stabilizers used, which is intended to improve weldability and likely has a minimal effect on the weld overlay mechanical performance (i.e. hardness and ASTM G65 testing).

The properties of the CFEXP alloys were measured using the below starting parameters, although slight variances occurred between welding individual alloys as described with respect to each figure. Each alloy was welded onto the joint in 3-4 consecutive slightly overlapping 1″ beads.

Substrate: 4137 Tool Joint 6⅝″ outer diameter

Pre-Heat=500° F.

Shielding Gas=98-2 (Argon/CO2) 45 CFH

Stick Out=1″

Wire Feed=4.5, Drag/Push Angle=5°

Voltage=29V, Amperage=310 A

Oscillation=50 Cycles/min

Rotation=1 min 48 s

Traverse Step=1⅛″

Overlap=⅛″

Interpass Temperature, 700° F. (temperature of joint in between subsequent weld beads)

CFEXP-1

FIGS. 25A and 25 B illustrate the result of welding the CFEXP-1 alloy onto a 6⅝″ 4137 steel tool joint with a single pass. The welding parameters were as follows: Pre-Heat=500° F., Shielding Gas=98-2 45 CFH, Stick Out=1″, Wire Feed=4.5, Drag/Push Angle=5°, Voltage=29V, Amperage=310 A, Oscillation=50 Cycles/min, Rotation=1 min 48 s, Traverse Step=1⅛″, Overlap=⅛″, Interpass Temperature, 700° F. FIG. 25 A illustrates a single bead and FIG. 25B illustrates four beads. In both cases, the weld was crack free.

CFEXP-2

FIGS. 26A and 26B illustrate single passes of as-welded CFEXP-2 alloy on 6⅝″ 4137 steel tool joint. The welding parameters were as follows: Pre-Heat=500° F., Shielding Gas=98-2 45 CFH, Stick Out=1″, Wire Feed=4.5, Drag/Push Angle=5°, Voltage=29V, Amperage=320 A, Oscillation=50 Cycles/min, Rotation=1 min 48 s, Traverse Step=1⅛″, Overlap=⅛″, Interpass Temperature, 715-745° F.

FIG. 26A illustrates a single bead and FIG. 26B illustrates four beads. In both cases, the weld was crack free.

CFEXP-5

FIG. 27 illustrates a single pass of as-welded CFEXP-5 alloy on 6⅝″ 4137 steel tool joint. The welding parameters were as follows: Pre-Heat=500° F., Shielding Gas=98-2 450 CFH, Stick Out=1″, Wire Feed=4.25, Drag/Push Angle=5°, Voltage=28.5V, Amperage=310-320 A, Oscillation=40 Cycles/min, Rotation=1 min 40 s, Traverse Step=1⅛″, Overlap=⅛″, Interpass Temperature, 700-720° F. The weld was found to be crack free.

CFEXP-6

FIGS. 28A and 28B illustrate single passes of as-welded CFEXP-6 alloy on 6⅝″ 4137 steel tool joint. FIG. 28A illustrates a single bead while FIG. 28B illustrates four beads. In both cases, the welds were found to be crack free. The welding parameters were as follows: Pre-Heat=500° F., Shielding Gas=98-2 45 CFH, Stick Out=1″, Wire Feed=4.5, Drag/Push Angle=5°, Voltage=28.5V, Amperage=300-310 A, Oscillation=40 Cycles/min, Rotation=1 min 48 s, Traverse Step=1⅛″, Overlap=⅛″, Interpass Temperature, 700-740° F.

CFEXP-11a

FIGS. 29A and 29B illustrate as-welded CFEXP-11a on 6⅝″ 4137 steel tool joint. FIG. 29A illustrates a single pass three bead weld and FIG. 29B illustrates a double pass three bead weld. In both cases, the welds were crack free. The welding parameters were as follows: Pre-Heat=500° F., Shielding Gas=98-2 40 CFH, Stick Out=1″, Wire Feed=4.5, Drag/Push Angle=5°, Voltage=28.5V, Amperage=300-310 A, Oscillation=40 Cycles/min, Rotation=1 min 48 s, Traverse Step=1⅛″, Overlap=⅛″,Interpass Temperature, 700-740° F.

The grain size of the ferritic (matrix) phase of the CFEXP-11b alloy when deposited onto a tool joint according to the described parameters above was determined via X-ray diffraction. X-ray diffraction is a standard method to determine the average grain size of materials. FIG. 35 shows the X-ray diffraction spectrum for the alloy and Table 3 shows the quantified peak parameters for the diffraction spectrum. Specifically, the X-ray diffraction technique was performed on the as-welded CFEXP-11b alloy sectioned from the single pass tool joint illustrated in FIG. 5A. Two phases could be identified using this technique, 1) ferritic iron which possess a slightly distorted lattice constant due to the presence of other soluble elements (Cr, Mo, W, . . . ), and 2) a iron carbide phase. Other phases such as Niobium carbide are likely present in the alloy but could not be identified to a low volume fraction. Based on the height to width ratios of the peaks corresponding to the ferritic iron peaks the average grain size was determined to be 16.1 nm.

TABLE 3 Quantified peak data for CFEXP-11b X-ray diffraction spectrum R = 7.33% Total Area = 69228 @ 2-Theta d(Å) Height Area(al) Area % FWHM XS(Å) 35.045 2.5584 19 1426 5.2 0.831 134 36.267 2.4750 24 776 2.8 0.841 132 42.705 2.1156 338 11512 41.9 0.740 162 44.507 2.0340 1179 27490 100.0 0.557 269 49.688 1.8334 91 4562 16.6 1.097 96 64.726 1.4391 118 10021 36.5 1.141 97 72.996 1.2951 42 3935 14.3 1.227 94 82.004 1.1741 198 9506 34.6 1.081 117

FIGS. 36A-36B are backscatter-mode scanning electron micrographs (SEMs) of the microstructure of the CFEXP-11 alloys. The microstructure is representative of all the Mo-containing alloys disclosed herein. Additionally, the microstructure is structurally similar to the W-containing alloys disclosed herein. FIG. 37 is a SEM of the microstructure of an example W-containing alloy—Fe (balance), Cr (5%), B (0.8%), C (0.97%), V (2%) Nb (4%), W (11.45%), Si (0.15%), Ti (0.25%) (in weight percent).

Both contain a fine-scale ferritic phase 10-20 nm in size (shown as the grey matrix phase 3603, 3703) with embedded Niobium carbide particles 1-10 μm in size (white precipitates 3601, 3701). The only difference between the Mo and W containing alloys is the compositions, although not morphology, of the darker grey phase 3602, 3702 which typically surrounds the Niobium carbide particles. This phase either possess a relatively higher concentration of Molybdenum or Tungsten in addition to chromium (similar to all CFEXP alloys). The energy dispersive spectroscopy for an alloy containing Mo and one containing W is shown in Table 4 and Table 5, respectively. As shown, both alloys are composed of a ferritic matrix with Niobium-rich phases, which have been identified as Niobium carbide particles via X-ray diffraction. The third phase, which is relatively richer in chromium and either Mo or W, has been characterized as ferritic iron in both alloy types via X-ray diffraction. In certain alloys, such as the example alloy shown in FIG. 37, additional hard precipitates such as complex W-borocarbides can precipitate. The formation of these Mo and/or W borocarbides is advantageous for increasing wear resistance. This may be desirable for single pass application but is considered undesirable in elevated volume fractions for a crack resistant alloy capable of double layer crack resistance on tool joints.

TABLE 4 Typical Energy Dispersive Spectroscopy for Mo-containing alloys Phase Fe Cr Nb Mo Ti Matrix balance 3.17 0 0.8 0 Niobium Carbide 6 1 >83 2-3 6 Cr-Enriched Matrix balance 10.25 0.6 4.4 0

TABLE 5 Typical Energy Dispersive Spectroscopy for W-containing alloys Phase Fe Cr Nb W Ti Matrix balance 3.4 0 3.4 0 Niobium Carbide 6 1 >80 4-5 5-6 Cr-Enriched Matrix balance 7.5 0 3.5 0

CFEXP-11 Testing Methods

The weld overlays were verified as crack-free initially through visual examination and then through either magnetic particle inspection or fluid dye penetrant testing. Coupons were sectioned from these samples (single pass) for use in hardness and ASTM G65 testing, and thus represent properties experienced in the field. In all cases, a second weld overlay pass made directly over the previous 3 band layer was attempted. Only a slight wire brush was used to clean the previous hardband layer from dust, no actual weld metal was removed in a significant way.

The results of the welding trials and mechanical testing are shown in Table 6. As shown, all of the experimental alloys can be successfully deposited crack free as a single layer weld onto the tool joint. In some applications it is desirable to have a thick weld layer between 8/32″ and 10/32″, which is typically achieved through controlling the welding parameters and applying a double pass overlay. It is furthermore, desirable to maintain a crack-free weld overlay at this thickness. As the results show, the CFEXP-11 and CFEXP-12 alloys could be deposited as double layer onto the tool joint without cracking. This unique attribute does not result in a loss in wear resistance, as these alloys (CFEXP-11 and CFEXP-12) also possess a ASTM G65 Procedure A mass loss of below 0.3 g. The ASTM G65 results for all the tested alloy of this disclosure are also plotted in FIG. 38. Typically, more ductile material can be welded as double pass layers without cracking, however, this is commonly accompanied by a decrease in hardness and/or wear resistance.

TABLE 6 Summary of CFEXP Alloy welding performance ASTM G65 Hardness Alloy # Single Pass Double Pass (g) (Rc) CFEXP-1 No cracks Cracking N/M N/M CFEXP-2 No cracks Cracking N/M N/M CFEXP-4 No cracks Cracking N/M N/M CFEXP-5 No cracks Cracking N/M N/M CFEXP-6 No cracks Cracking N/M N/M CFEXP-7 No cracks Cracking N/M N/M CFEXP-11a No cracks No cracks 0.183 58 CFEXP-12 No cracks No cracks 0.261 58 CFEXP-13 No cracks Cracking 0.326 56 CFEXP-14 No cracks Cracking 0.198 58-59 CFEXP-15 No cracks Cracking N/M N/M

The ability to be deposited as a double layer crack free overlay is not inherent in the general compositional range of these alloys or the fine-grained microstructure. To verify that the unique and unexpected properties of the CFEXP-11 alloy were not artifacts of optimal manufacturing or testing conditions, the chemistry was remade and subject to an additional round of testing. Two additional CFEXP 11 manufacturing variants were produced: CFEXP-11b (6) and CFEXP-11b (7). The pictures from the welding trials are shown in FIGS. 34A and 34B, where FIG. 34A illustrates the results of welding with CFEXP-11b(7) and FIG. 34B illustrates the results of welding with CFEXP-11b(6). The alloys demonstrated no cracking in two pass weld overlays to achieve a total weld thickness of 8/32″ to 10/32″, respectively. In these trials, the variants were welded onto 6⅝″ 4137 steel tool joints. The welding parameters were as follows: Pre-Heat=510° F., Shielding Gas=98-2 37 CFH, Stick Out=1″, Wire Feed=N/M, Drag/Push Angle=5°, Voltage=29V, Amperage=295-300 A, Oscillation=70 Cycles/min, Rotation=2 min 50 s, Traverse Step=1⅛″, Overlap=⅛″, Interpass Temperature, 630-670° F.

Coupons were cut from single pass overlays of these two alloys [CFEXP-11b (6) and CFEXP-11 (7)] and ASTM G65 Procedure A testing was conducted as shown in Table 7. As shown, this alloy chemistry maintains a high hardness with corresponding high wear resistance as well as the ability to be welded as a double layer onto a 6⅝″ tool joint without cracking.

TABLE 7 Details of single pass weld overlay CFEXP-11b wear and hardness testing Alloy # ASTM G65 Hardness Facility CFEXP-11b (6) 0.216 60 1 CFEXP-11b (6) 0.216 59 1 CFEXP-11b (7) 0.218 59 1 CFEXP-11b (7) 0.233 60 1 CFEXP-11b (6) 0.1943 N/M 2 CFEXP-11b (6) 0.1859 N/M 2 CFEXP-11b (7) 0.2035 N/M 2 CFEXP-11b (7) 0.2121 N/M 2 CFEXP-11b (6) 0.1608 58.5 3 CFEXP-11b (6) 0.1711 58.5 3 CFEXP-11b (7) 0.1725 57.5 3 CFEXP-11b (7) 0.1933 57.25 3 AVERAGE 0.198 58.72 N/A STDEV 0.022 1.0 N/A

FIGS. 30A and 30B illustrate as-welded CFEXP-12 alloy on 6⅝″ steel pipe indicating. FIG. 30A illustrates a single pass and FIG. 30B illustrates a double pass. In both cases, the weld was crack free. The welding parameters were as follows: Pre-Heat=500° F., Shielding Gas=98-2 45 CFH, Stick Out=1″, Wire Feed=4.5, Drag/Push Angle=5°, Voltage=29V, Amperage=320 A, Oscillation=50 Cycles/min, Rotation=1 min 48 s, Traverse Step=1⅛″, Overlap=⅛″, Interpass Temperature, 715-745° F.

CFEXP-13

FIGS. 31A and 31B illustrate as welded CFEXP-13 alloy on 6⅝″ steel pipe. FIG. 31A illustrates a single pass and FIG. 31B illustrates a double pass. In both cases, the weld was crack free. The welding parameters were as follows: Pre-Heat=500° F., Shielding Gas=98-2 45 CFH, Stick Out=1″, Wire Feed=4.5, Drag/Push Angle=5°, Voltage=29V, Amperage=320 A, Oscillation=50 Cycles/min, Rotation=1 min 48 s, Traverse Step=1⅛″, Overlap=⅛″, Interpass Temperature, 715-745° F.

CFEXP-14

FIGS. 32A-C illustrate as-welded CFEXP-14 alloy on 6⅝″ 4137 steel tool joint. FIG. 32A illustrates a single pass weld overlay and was found to be crack free. FIG. 32B illustrates a double pass weld overlay and was found to contain a crack 3200, illustrated in FIG. 32C. The welding parameters were as follows: Pre-Heat=500° F., Shielding Gas=98-2 45 CFH, Stick Out=1″, Wire Feed=4.5, Drag/Push Angle=5°, Voltage=29V, Amperage=320 A, Oscillation=50 Cycles/min, Rotation=1 min 48 s, Traverse Step=1⅛″, Overlap=⅛″, Interpass Temperature, 715-745° F.

CFEXP-15

FIG. 33 illustrates as-welded CFEXP-15 alloy on 6⅝″ 4137 steel tool joint indicating no cracks. The welding parameters were as follows: Pre-Heat=500° F., Shielding Gas=98-2 45 CFH, Stick Out=1″, Wire Feed=4.5, Drag/Push Angle=5°, Voltage=29V, Amperage=320 A, Oscillation=50 Cycles/min, Rotation=1 min 48 s, Traverse Step=1⅛″, Overlap=⅛″, Interpass Temperature, 715-745° F.

Alloy Group CrF

Some embodiments of the invention comprises a composition of matter in the following range:: a balance of Fe; between 3-5 wt. % Nb; between 0-2 wt. % V; between 0.75-2 wt. % C; between 0.5-2 wt. % B; between 10-11.45 wt. % W; between 0.1-0.3 wt. % Ti; and between 0.1-0.4 wt. % Si. For example, these compositions can be alloys, welds, or welding wires. In some applications it is desirable to have alloys which do not have any chromium content. One reason for this desired metallurgy is to prevent the production of hexavalent chromium fumes, a known carcinogen, during welding. The alloys disclosed here do not rely on the formation of chromium containing carbides or borides to exhibit the desired properties such as high hardness or wear resistance. To demonstrate this, several alloys with similar chemistries, except for the lack of chromium were produced in alloy ingot form. Measured hardness values for these alloys, labeled as CrF (‘chromium-free’) variants were measured and are shown in Table 8, and range from 50 Rc to above 60 Rc. The CrF-6 alloy was selected for manufacture into a cored wire for welding trials, and due to manufacturing tolerances the CrF-7 chemistry was produced. Welding trials on flat steel panels showed that this chemistry produced a 50-55 Rc layer in the as-welded condition.

TABLE 8 Summary of CrF cast alloy performance Hardness Alloy # (Rc) CrF-3 53-55 CrF-4 52-54 CrF-5 59-61 CrF-6 53-55 CrF-7 50-55

While various embodiments of the present invention have been described above, it should be understood that they have been presented by way of example only, and not of limitation. Likewise, the various diagrams may depict an example architectural or other configuration for the invention, which is done to aid in understanding the features and functionality that can be included in the invention. The invention is not restricted to the illustrated example architectures or configurations, but the desired features can be implemented using a variety of alternative architectures and configurations. Indeed, it will be apparent to one of skill in the art how alternative functional, logical or physical partitioning and configurations can be implemented to implement the desired features of the present invention. Also, a multitude of different constituent module names other than those depicted herein can be applied to the various partitions. Additionally, with regard to flow diagrams, operational descriptions and method claims, the order in which the steps are presented herein shall not mandate that various embodiments be implemented to perform the recited functionality in the same order unless the context dictates otherwise.

Although the invention is described above in terms of various exemplary embodiments and implementations, it should be understood that the various features, aspects and functionality described in one or more of the individual embodiments are not limited in their applicability to the particular embodiment with which they are described, but instead can be applied, alone or in various combinations, to one or more of the other embodiments of the invention, whether or not such embodiments are described and whether or not such features are presented as being a part of a described embodiment. Thus, the breadth and scope of the present invention should not be limited by any of the above-described exemplary embodiments.

Terms and phrases used in this document, and variations thereof, unless otherwise expressly stated, should be construed as open ended as opposed to limiting. As examples of the foregoing: the term “including” should be read as meaning “including, without limitation” or the like; the term “example” is used to provide exemplary instances of the item in discussion, not an exhaustive or limiting list thereof; the terms “a” or “an” should be read as meaning “at least one,” “one or more” or the like; and adjectives such as “conventional,” “traditional,” “normal,” “standard,” “known” and terms of similar meaning should not be construed as limiting the item described to a given time period or to an item available as of a given time, but instead should be read to encompass conventional, traditional, normal, or standard technologies that may be available or known now or at any time in the future. Likewise, where this document refers to technologies that would be apparent or known to one of ordinary skill in the art, such technologies encompass those apparent or known to the skilled artisan now or at any time in the future.

The presence of broadening words and phrases such as “one or more,” “at least,” “but not limited to” or other like phrases in some instances shall not be read to mean that the narrower case is intended or required in instances where such broadening phrases may be absent. The use of the term “module” does not imply that the components or functionality described or claimed as part of the module are all configured in a common package. Indeed, any or all of the various components of a module, whether control logic or other components, can be combined in a single package or separately maintained and can further be distributed in multiple groupings or packages or across multiple locations.

Additionally, the various embodiments set forth herein are described in terms of exemplary block diagrams, flow charts and other illustrations. As will become apparent to one of ordinary skill in the art after reading this document, the illustrated embodiments and their various alternatives can be implemented without confinement to the illustrated examples. For example, block diagrams and their accompanying description should not be construed as mandating a particular architecture or configuration. 

1-23. (canceled)
 24. A composition of matter comprising: Fe; between 4-6 wt. % Cr; between 0.8-1.2 wt. % Mn; between 4-5 wt. % Nb; between 0-1 wt. % V; between 0.6-1.1 wt. % C; between 0.1-0.5 wt. % Ti; and between 0.4-0.75 wt. % Si.
 25. The composition of matter of claim 24, further comprising: B in an amount of 2.25 wt. % or less; and Mo in an amount of 4 wt. % or less.
 26. The composition of matter of claim 24, wherein the composition is a welding wire.
 27. The composition of matter of claim 24, wherein the composition is a weld.
 28. An alloy comprising: Fe; between 4-6 wt. % Cr; between 0.8-1.2 wt. % Mn; between 4-5 wt. % Nb; between 0-1 wt. % V; between 0.6-1.1 wt. % C; between 0.1-0.5 wt. % Ti; and between 0.4-0.75 wt. % Si.
 29. The alloy of claim 28, further comprising: B in an amount of 2.25 wt. % or less; and Mo in an amount of 4 wt. % or less.
 30. The alloy of claim 28, wherein the alloy has a Rockwell C hardness greater than
 50. 31. The alloy of claim 30, wherein the alloy has a Rockwell C hardness greater than
 55. 32. The alloy of claim 28, wherein the alloy has a microstructure comprising a fine-grained matrix, wherein the matrix comprises Nb-carbide precipitates having sizes less than 10 μm and hard precipitates having grain sizes less than 10 μm.
 33. The alloy of claim 28, wherein the alloy is capable of being deposited as a weld overlay coating.
 34. The alloy of claim 28, wherein the alloy is capable of being deposited using a MIG welding technique on a tool joint.
 35. The alloy of claim 28, wherein the alloy is capable of being deposited crack-free when deposited on a substrate that is pre-heated to at least 500° F.
 36. The alloy of claim 28, wherein the alloy is capable of being welded in two layers onto a 4137 6⅝″ O.D. tool joint to achieve a total weld thickness of at least 8/32″ without cracking.
 37. The alloy of claim 36, wherein the alloy is capable of being deposited as a 10/32″ thick double pass weld overlay without cracking.
 38. The alloy of claim 36, wherein the alloy exhibits a mass loss less than 0.3 g lost in ASTM G65 Procedure A. 